Method for casting

Abstract

A method for casting that includes a.) determining a diameter (D) of a cross section of a product to be cast in meter (m), b.) determining an intended steady-state casting speed (V) of the product to be cast using direct chill casting in meter per second (m/s), c.) determining a Si content (cSi) in percent by weight based on the total weight of a melt (wt-%) for the melt to be used for casting the cast product, d.) preparing a melt comprising Zn: 5.30 to 5.9 wt-%, Mg: 2.07 to 3.3 wt-%, Cu: 1.2 to 1.45 wt-%, Fe: 0 to 0.5 wt-%, Si: according to cSi, impurities up to 0.2 wt-% each and 0.5 wt-% in total, and balance aluminium, and e.) casting the melt into the cast product having the intended diameter (D) using direct chill casting, wherein the casting is carried out using the intended steady-state casting speed (V).

Claims

1. A method for casting comprising a.) determining a diameter (D) of a cross section of a product to be cast in meter (m), b.) determining an intended steady-state casting speed (V) of the product to be cast using direct chill casting in meter per second (m/s), c.) determining a Si content (cSi) in percent by weight based on the total weight of a melt (wt-%) for the melt to be used for casting the cast product, wherein the intended diameter (D), the intended steady-state casting speed (V) and the intended Si content (cSi) are determined such that the equations
V*D≤0.00057−0.0017*cSi  (I)
and
V*D≥0.00047−0.0017*cSi  (II)
and
cSi≤0.1  (III) are fulfilled, d.) preparing a melt comprising Zn: 5.30 to 5.9 wt-%, Mg: 2.07 to 3.3 wt-%, Cu: 1.2 to 1.45 wt-%, Fe: 0 to 0.5 wt-%, Si: according to cSi, impurities up to 0.2 wt-% each and 0.5 wt-% in total, and balance aluminium, e.) casting the melt into the cast product having the intended diameter (D) using direct chill casting, wherein the casting is carried out using the intended steady-state casting speed (V).

2. The method according to claim 1, wherein two out of the three variables V, D and cSi are determined based on product or process requirements and the third variable is calculated using equations (I) to (III).

3. The method according to claim 1, wherein the casting the melt into the cast product is carried out using between 14 and 20 cubic meter per hour and meter of intended diameter (m3/(h*D)) cooling water for the direct chill casting.

4. The method according to claim 1, wherein in the preparing the melt, between 0.025 and 0.1 wt-% grain refiner based on Al, Ti and/or B are added to the melt.

5. The method according to claim 1, wherein the diameter (D) of the product to be cast is the largest circle equivalent diameter in a cross section of the product to be cast.

6. The method according to claim 1, wherein the diameter (D) of the product to be cast is larger than 450 mm and wherein optionally a wiper is used to remove water from the casted product, and wherein optionally the wiper is arranged such that it is on a vertical level of a bottom of the solidification zone of the product during steady-state casting.

Description

SHORT DESCRIPTION OF THE FIGURES

(1) FIG. 1 shows calculated evolutions of solid fractions for alloys according to the invention and according to a comparative example with different Fe and Si contents.

(2) FIG. 2 shows a direct chill casting mold schematically in a horizontal cross section.

(3) FIG. 3 shows temperature field in view (a), accumulated volumetric strain in view (b) and integrated critical strain in view (c) for alloy A2 at a casting length of approx. 1 m.

(4) FIG. 4 shows mean stress in view (a), peak principal stress in view (b) and critical cracking size in view (c) for alloy A2 at a casting length of approx. 1 m.

(5) FIG. 5 shows the integrated critical strain from bottom to top through the center of a cast product, here a cylindrical billet, for alloys A2, A3, A6 and A7.

(6) FIG. 6 shows the process window for casting depending on Si content (cSi), casting speed and diameter of the cast product according to embodiments of the present invention.

DETAILED DESCRIPTION OF THE INVENTION

(7) Numerical simulations as well as industrial trials were carried out. The computer simulations involve microstructure simulations as well as casting process simulations. The industrial trials involve casting of billets (generally cylindrical cast products) having a diameter of 405 mm with varying chemical compositions. The billets were cast using a casting system as described e.g. in European Patent Specification EP1648635B1, which is incorporated herein by reference, or in A. Hakonsen, J. E. Hafsas, R. Ledal, Light Metals, TMS, San Diego, Calif., USA, 2014, 873-878.

(8) Numerical Simulations

(9) The numerical simulations involved the development of models that were then, in combination with appropriate data as described below, used for simulations to confirm the effectiveness of the embodiments of the present invention.

(10) Microstructure Model

(11) The Scheil model coded in the software Thermo-Calc (Version S by Thermo-Calc Software AB, Solna, Sweden) together with the TTAL7 database (developed by Thermotech Ltd., available via Thermo-Calc Software AB) has been used to calculate the solidification paths. The Scheil model is not able to predict how the cooling rate influences the microstructure formation. It is built on the assumptions that no diffusion occurs in the solid and that there is complete mixing in the liquid during solidification. Therefore, only the effect of alloy chemistry on the solidification path evolution is considered, while this model ignores kinetic factors such as diffusion.

(12) Process Model

(13) The Alsim model (e.g. described in D. Mortensen: Metallurgical and Materials Transactions B, 1999, 30B, 119-133. H. G. Fær and A. Mo: Metallurgical Transactions B, 1990, 21B, 1049-1061 and H. J. Thevik, A. Mo and T. Rusten: Metallurgical and Materials Transactions B, 1999, 30B, 135-142) is a finite element model for transient simulations of heat, fluid flow, macrosegregation, stresses and deformation for continuous casting processes. For direct chill (DC) casting, boundary conditions are described with a very high level of details regarding contact zones, air gap sizes, and water hitting points. The effects of stresses and displacements on contact zones, i.e. air gap formation between ingot and mould or bottom block, are accounted for in the thermal boundary conditions. Transient temperature and fraction of solid fields are input to a two-phase mechanical model presented in detail in the article: H. J. Thevik, A. Mo and T. Rusten: Metallurgical and Materials Transactions B, 1999, 30B, 135-142. The mechanical analysis is carried out both in the fully solid regions of the ingot as well as in the coherent part of the mushy zone. The upper boundary of the coherent mushy zone corresponds to the solid volume fraction at coherency that is input to the model. The hot cracking susceptibility is estimated by the integrated critical strain (ICS) as further described e.g. in M. M'Hamdi, A. Mo, H. G. Fjær, Metallurgical and Materials Transactions A, 2006, 37, 3069. The criterion is taking into account both the lack of melt feeding during solidification and thermal deformation, as these two phenomena are the main driving forces for hot tearing during DC casting:

(14) $\begin{array}{cc}\mathrm{\Delta .Math.}\left(w_v,w_d\right)=\{\begin{array}{c}0\\ t(g_s=g_s^{\mathrm{nof}}\\ \int \\ t\left(p_1<p_c\right)\end{array}\left(w_v.Math.\mathrm{tr}\left({\stackrel{.}{\mathrm{.Math.}}}_s^p\right)+w_d.Math.{\stackrel{\stackrel{\_}{.}}{\mathrm{.Math.}}}_s^p\right)\mathrm{dt}\begin{array}{c}\mathrm{for}{p}_1<p_c\\ \mathrm{for}{p}_1<p_c\end{array}& \left(1\right)\end{array}$
This hot cracking indicator ensures that no hot cracking occurs without insufficient feeding. This is taken care of by introducing a critical liquid pressure drop, pc. Above this value it is assumed that liquid feeding will prevent the formation of hot cracks even in the presence of a tensile stress state. When the pressure drop is lower than the critical value, volumetric and deviatoric viscoplastic (weighted by the functions wv and wd) straining of the material are assumed to contribute to the widening of existing pores and their growth into hot cracks. The parameter “gsnof” denotes the solid fraction at which coalescence and bridging between the grains in the microstructure of the cast product are fairly advanced and the alloy has obtained sufficient ductility to prevent the formation of a hot crack.

(15) For cold cracking, the cracking susceptibility is estimated using a critical crack size (CCS) criterion as described in detail e.g. in the article: M. Lalpoor, D. G. Eskin, L. Katgerman, Metallurgical and Materials Transactions A, 2010, 41, 2425. The principle idea of the criterion is that if the defect size (i.e. a hot crack) exceeds the CCS at temperatures when the material is brittle, cold cracking will occur. The criterion accounts for the geometry of the initial defect (e.g. penny-shaped or thumbnail-shaped) as well as the temperature dependent plane strain fracture toughness (Klc). For example, for a penny-shaped (volumetric) crack the criterion is given by:

(16) $\begin{array}{cc}{a}_c=\frac{\pi }{4}{\left(\frac{K_{Ic}}{{\sigma }_{11}}\right)}^2& \left(2\right)\end{array}$
where σ11 is the first principal stress σ11.
Microstructure Simulations

(17) A series of simulations have been carried out for the alloys listed in Table 1 to simulate how variations in alloying content influence the solidification path and the phase formation towards the end of solidification. The alloying components, Zn, Mg, and Cu are kept fixed while the alloying components Fe and Si are added with different ratios.

(18) FIG. 1 shows the last part of solidification for the alloys with varying Fe and Si content. That is, FIG. 1 shows the calculated evolutions of solid fraction for the model alloys A1 to A7 as shown in Table 1 with different Fe and Si contents.

(19) It is apparent that the alloys with the highest Si content has a wider solidification interval by 15° C. The reaction which terminates the solidification for the alloys with low Si is
Liquid.fwdarw.Mg2Si+MgZn2  (3)
where the MgZn2 phase also contains Cu, i.e. the phase composition is 33 at % Mg, 30 at % Cu, 16 at % Zn and 11 at % Al. Increasing the Si content leads to a longer solidification interval as Si reacts with Mg to form Mg2Si. Less Mg will then be available for formation of the MgZn2-phase. If the amount of MgZn2 phase is insufficient to tie up all the Cu in liquid solution, low melting Cu containing phases, e.g. Al2CuMg_S and Al7Cu2M will form resulting in a wider solidification range. The iron bearing phases, are early forming phases and the variations in Fe are found to have no influence on the end of solidification and the solidification interval length.

(20) TABLE-US-00001 TABLE 1 Composition of model alloys in wt-% with balance aluminium Alloy Zn Mg Cu Fe Si A1 5.85 2.3 1.4 0.7 0.1 (comparative) A2 0.2 0.1 A3 0.3 0.15 A4 0.1 0.1 A5 0.2 0.2 A6 0.1 0.2 A7 0.15 0.3
Process Simulations

(21) Cracking tendencies of the model alloys A2, A3, A6 and A7 have been compared by process modelling. Fully coupled heat transfer, flow and mechanical simulations were performed for casting of billets of the model alloys with diameter 405 mm using the LPC casting technology as described e.g. in EP1648635B1. The 2D axis-symmetric start up geometry and mesh is shown in FIG. 2. The solidification paths from ThermoCalc and thermophysical properties, e.g. densities, thermal conductivity, heat capacity and heat of fusion as function of temperature, calculated using the Alstruc software (see e.g. A. L. Dons. E. K. Jensen. Y. Langsrud. E. Tromborg and S. Brusethaug: Metallurgical and Materials Transactions A. 1999. 30A. 2135-2146) were used as input to the thermal model. For the constitutive mechanical equations, mushy zone parameters were extracted from the experimental 7050 data published in T. Subroto, A. Miroux, D. G. Eskin, K. Ellingsen, A. Marson, M. M'Hamdi and L. Katgerman, Proc. 13th International Conference on Fracture, Beijing, China, 2013, 9. For the fully solidified solid, the 7050 data published in M. Lalpoor, D. G. Eskin, and L. Katgerman, Materials Science and Engineering A, 2010, 527; 1828-1834 was used. The mechanical data used as input to the model are the same for all alloys and only the effect of the alloy chemistry on the solidification path and thermophysical properties are taken into account.

(22) Transient simulations were performed until a casting length of 1 meter was reached. For all experiments, the casting speed was ramped up from 30 to 36 mm/min (millimeter per minute) after a short holding period of 30 s seconds and then kept constant (steady-state casting speed). The water amount was set to 7 m3/h (cubic meter per hour).

(23) FIG. 2 shows the 2D start geometry and mesh. During casting, the melt is led into the mold via a melt inlet. In the mold, the melt is cooled using cooling water. The bottom or starter block is moved vertically downwards while melt flows continuously into the mold to produce the cast product. The speed, with which the bottom block is moved vertically downwards, is referred to as the casting speed. A casting speed that is too high will result in a cast product having cracks. A casting speed that is too low will result in a poor utilization of the casting equipment and a low production amount over time.

(24) FIG. 3 shows the temperature field, the accumulated volumetric strain as well as the integrated critical strain (ICS) after a casting length of 1 m for alloy A2. View (a) of FIG. 3 shows the temperature field, view (b) shows the accumulated volumetric strain and view (C) shows the integrated critical strain. As is apparent e.g. from FIG. 3, the highest ICS values are found in the billet centre and the start-up period was found to be the most relevant phase for formation of centre cracks.

(25) The critical crack size criterion is shown together with the peak principal stress and the mean stress for alloy A2 in FIG. 4. The mean stress field shown in view (a) of FIG. 4 reveals compressive stresses at the surface and tensile stresses in the centre. The highest stress values in any direction as seen by the peak principal stress field (120 MPa) shown in view (b) of FIG. 4 are found in the center in the lower part of the casting. The areas with the smallest critical crack size are found in the same areas and the model indicates that defects in the order of 5 mm would propagate as cold cracks. The areas with the highest hot cracking sensitivity is coinciding with the areas with the smallest critical crack size and could be potential initiation points for cold cracking as is e.g. apparent from view (c) of FIG. 4.

(26) FIG. 5 shows values for the integrated critical strain through the billet center for all four alloys A2, A3, A6 and A7. The ranking of the hot cracking tendency follows the solidification interval length. The liquid pressure drop is found to be significantly higher indicating a more difficult liquid feeding of the mushy zone for the longer solidification intervals leading to a higher ICS value. As an increase in the Si content leads to longer solidification intervals, the hot cracking tendency correlates with the Si content.

(27) Physical Experiments

(28) A series of billets with varying chemical compositions as given in Table 2 were produced using direct chill casting as described in EP1648635B1, which is incorporated herein by this reference. Generally speaking and with reference to FIG. 2, a direct chill casting mold has openings on the top and the bottom. The melt is introduced into the mold via the top opening, at least partially solidifies in the mold to form the cast product. To facilitate solidification, water cooling may be used. Water may be led through water jackets in the mold and is sprayed on the at least partially solidified cast product exiting the mold. The total amount of water used during casting influences the cooling rate of the cast product. The cast product exits the mold via the bottom opening while it is supported on the downwards moving bottom block. The speed with which the cast product exists the mold is referred to as the casting speed or vertical casting speed. Herein, the casting speed refers to the steady state phase after the starting phase of a casting operation. The casting speed mentioned in the patent claims may be the maximum casting speed during the total casting operation (from startup phase to end of casting) according to the invention.

(29) TABLE-US-00002 TABLE 2 Composition of experimental alloys in wt-%, balance aluminium, and casting speed in mm/min at which cracking occurs. Cast # Fe Si Mg Zn Cu V.sub.critical 1 0.19 0.06 2.68 5.54 1.34 67.5 2 0.25 0.12 2.62 5.34 1.25 59 3 0.22 0.14 2.47 5.49 1.36 57.6 4 0.47 0.14 2.31 5.4 1.43 57 5 0.27 0.14 2.49 5.53 1.4 41.5 6 0.28 0.14 2.39 5.48 1.42 36 7 0.28 0.14 2.39 5.48 1.42 49 8 0.4 0.2 2.07 5.47 1.37 36 9 0.23 0.21 2.5 5.72 1.5 36 10 0.23 0.21 2.5 5.72 1.5 35 11 0.1 0.23 2.76 5.68 1.47 35 12 0.1 0.23 2.76 5.68 1.47 36 13 0.11 0.24 3.29 5.47 1.42 39 14 0.11 0.25 2.68 5.61 1.39 48 15 0.1 0.25 3.05 5.67 1.45 36 16 0.41 0.4 2.1 5.66 1.47 33.9

(30) Six billets were cast in parallel for the present experiments. The cooling conditions were kept similar for all castings. After reaching the steady state, the casting speed was slowly ramped up until cold cracking in two billets occurred. The casting speed when two billets had a cold crack is denoted “critical casting speed” (V.sub.Critical) and is given in millimeter per minute. The cold cracking was observed through the audible sound when the cold crack was forming. It was found that the alloys with higher Si content cracked at lower casting speeds, whereas the alloys with a low Si content cracked at higher casting speeds or did not crack. The correlation between the Si content and the critical casting speed is shown in FIG. 6. The observed behavior is explained by longer solidification intervals due to formation of low-melting phases resulting in increasing cracking tendency in the billet center as is also confirmed by the numerical simulations. It is also confirmed by the numerical simulations together with the mechanism of heat transfer, that the diameter of the cast product has an influence on the critical casting speed. It is further found from heat transfer considerations that the diameter of a cast product can be approximated as the largest circle equivalent diameter of a cast product in a—with respect to the vertical casting direction—horizontal cross section of the cast product.

(31) The inventors found that the critical casting speed is generally independent of the content of Mg, Cu, Fe, and Zn of the melt. The inventors also found that the critical casting speed and the Fe/Si-ratio are independent from each other. However, to improve casting efficiency and product properties, the alloy used in the method according to the present invention may optionally comprise a minimum of 0.01 wt-% Si.

(32) Accordingly, to achieve efficient casting and to produce an efficient cast product, the contents of Mg, Cu, Fe and Zn may be chosen based on desired product properties. However, to ensure good mechanical properties and corrosion resistance of the cast product, Zn is limited to 5.30 to 5.9 wt-%, Mg is limited to 2.07 to 3.3 wt-%, Cu is limited to 1.2 to 1.45 wt-%, and Fe is limited to 0 to 0.5 wt-%. According to embodiments, the Zn content may be limited to 5.60 to 5.80 wt-%. According to embodiments, the Mg content may be limited to 2.30 to 2.50 wt-%. According to embodiments, the Cu content may be limited to 1.20 to 1.40 wt-%. Said narrower limits for Zn, Mg and/or Cu may give the cast product better mechanical properties and corrosion resistance while the tendency to form cracks remains low when the casting is carried out according to the present invention. According to the invention, the balance is aluminium. Impurities may be included in the alloy according to the invention up to 0.20 wt-% for each element and up to 0.50 wt-% in total.

(33) When the casting conditions in direct chill casting for such an alloy do not fulfill equation V*D≤0.00057−0.0017*cSi, wherein V is the casting speed (that is the vertical speed of the bottom block) in meter per second, D is the diameter (for example the largest circle equivalent diameter in meter) of the cast product in meter and cSi the silicon content of the alloy in weight percent, cracking occurs resulting in a cast product with poor quality. On the other hand, when the casting conditions do not fulfill equation V*D≥0.00047−0.0017*cSi, then there is no efficient use of the casting equipment and the production rate of the cast product is insufficient.

(34) When the silicon content of the melt, cSi, is higher than 0.1 wt-%, (and consequently also the silicon content of the alloy that forms the cast product after solidification of the melt), the mechanical product properties deteriorate and in addition the alloy/melt requires a casting speed that is too low.

(35) Accordingly, as shown in FIG. 6, the Si content may be chosen based on the desired casting speed to allow efficient use of the casting equipment, or, if the Si content is fixed due to product specification, an optimal casting speed may be chosen. When the process window according to the present invention is used, the casting process can be optimized to cast alloys of the AA7xxx type with the highest possible speed while maintaining product quality.